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An active tendon, consisting of a displacement actuator and a co-located force sensor, has been adopted by many studies to suppress the vibration of large space flexible structures. The damping, provided by the force feedback control algorithm in these studies, is small and can increase, especially for tendons with low axial stiffness. This study introduces an improved force feedback algorithm, which is based on the idea of velocity feedback. The algorithm provides a large damping ratio for space flexible structures and does not require a structure model. The effectiveness of the algorithm is demonstrated on a structure similar to JPL-MPI. The results show that large damping can be achieved for the vibration control of large space structures.

In general, large flexible space structures contain cable elements [1]. The cables are adopted to increase the stiffness of flexible structures, to maintain structure configuration, and to eliminate geometric uncertainty due to gaps. In recent years, a further step in exploiting the potential of cables has been proposed, whereby the cable acts as an active tendon to suppress structural vibrations. The idea was first presented for the vibration attenuation of bridges and buildings [2]. Researchers have introduced a lot of control algorithms for the active tendon. Leipholz and Abdel-Rohman [2] adopted a pole assignment method and optimal control method to attenuate the vibration of bridges and buildings. Betti and Panariello [3] adopted a linear quadratic regulator (LQR) to suppress the vibration of a building with a single degree of freedom (DOF). Chuang and Wu [4] extended the LQR to buildings with multi-DOFs to avoid structure destruction. Chang and Yu [5] proposed an optimal pole placement technique for the vibration control of a structure under a white noise ground excitation. Agrawal and Yang [6] investigated the performance of an optimal polynomial control method for the vibration suppression of a benchmark problem. Bani-Hani et al. [7] used a neural network control method for experimental vibration attenuation of a 1/4 scale model of a three-story steel frame. Kim and Yun [8] presented a sliding mode fuzzy control (SMFC) algorithm for vibration reduction of large structures. Lin et al. [9] adopted Hinfinity optimality and H2 optimality to control the vibration of buildings with the soil-structure interaction (SSI) effect. Nudehi et al. [10] explored the use of end forces for vibration control in a cantilever beam with unilateral saturated nonlinear tendons. Then, Issa et al. [11] adopted this nonlinear tendon for vibration suppression in space structures.

Most control schemes are based on an accurate model of the structure. However, when the model of the structure is not precisely defined or some active tendons fail, the performance of those control schemes deteriorates and can even cause instability of the control system. As a result, some studies have adopted decentralized schemes, which consist of independent controllers to activate specific tendons with only local feedback information. The decentralized schemes are useful for high dimensional large space structures, and can also be adapted to address the failure of some active tendons. Magana et al. [12] introduced a robust decentralized active control scheme based on the Lyapunov stability approach. Cao et al. [13] proposed a set of decentralized controllers that minimize the performance index of each subsystem to control the vibration of cable-stayed bridges subjected to vertical seismic excitation, Luo et al. [14] adopted a sliding mode decentralized controller to reduce structure vibrations by considering uncertainties in the parameters of stay cable geometry and unknown environmental excitation. Xu and Wu [15] proposed a decentralized non-parametric identification and control strategy with artificial neural networks for large-scale structures by using a neural network control scheme to reduce structure vibrations. Overall, these control schemes are complex and difficult to realize in practice. Preumont and colleagues [16–18] proposed an active tendon and integral force feedback algorithm to attenuate structure vibrations. The active tendon consists of a displacement actuator (piezoelectric actuator) and a co-located force sensor on the cable end. The preloaded active tendon is installed on the structure, as shown in Figure 1. By measuring the tension change T and controlling the active displacement, the vibration can be suppressed. The integral force feedback control algorithm is:
(1)u=−gTswhere g is the integral feedback coefficient, u is the active displacement, and
1s is the integral operator. Guo et al. [19] added a proportionality factor to the feedback law of Equation (1) and presented a proportional-integral (PI) algorithm to improve control effectiveness. The two control algorithms do not depend on the space structure model, and they are stable for the controlled structure. The control algorithm is simple, and the effectiveness of the algorithm is high. However, the achievable maximal damping ratio can be increased, especially for tendons with low axial stiffness.

This study presents a differential force feedback algorithm to suppress structure vibrations. The algorithm can introduce large active damping to structures. The kernel idea of the control algorithm is velocity feedback, so the stability of the control system can be guaranteed. The control algorithm is simple, and also, no structural model is required.

The paper is organized as follows: in Section 2, the governing equation of the structure is presented and the differential force feedback strategy is addressed. In Section 3, the stability and effectiveness of the control algorithm are discussed for when there are discrepancies between the actual axial stiffness of the tendon and the stiffness used for control law design. In Section 4, a simulation is demonstrated on a free-free structure similar to JPL-MPI [18], and the effectiveness of the control algorithm is investigated. Conclusions are drawn in Section 5.

2.Control Strategy

The mass of an active tendon in a large space structure is usually small compared with the mass of the truss structure. As a result, the dynamics of the active tendon can be restricted to the tension in the tendon in the vibration control and its interaction with the structure. A multi-tendon system is considered in the following deduction, where the number of tendons is n. The governing equation for the structure is:
(2)Ms2x+Kx=∑i=1nbiTiwhere M and K denote the structure mass and stiffness matrices without active tendons; Ti is the tension on the ith tendon, and bi is the influence matrix of the ith tendon. The amount of damping on the large space structure is low, so it is neglected in the equation. Here, the mass of the tendon is small and neglected in the governing equation [16], therefore, the tendon can be considered as a spring. The tension in the ith tendon is derived from the structure vibration and the tip displacement of the active tendon as follows:
(3)Ti=kci(ui−biTx),i=1,2,⋯,nwhere kci is the stiffness of the ith active tendon, biTx is the relative displacement between the installation location of the ith tendon on the space structure; and ui is the active displacement. Since the displacement actuator and the force sensor are co-located, the influence matrix bi is identical in Equations (2) and (3).

The control algorithm is the differential force feedback:
(4)ui=kfi(sTi−kcisui),i=1,2,⋯,nwhere kfi is the feedback coefficient of the ith active tendon. After eliminating the tension caused by the active displacement, the residual tension on the tendon is proportional to the vibration displacement. Therefore, the active displacement in Equation (4) is proportional to the velocity of the installation locations of the tendon, and the control algorithm increases the amount of damping to the structure. All controllable and observable states are asymptotically stable. From Equation (4), the active displacements of the ith tendon can be expressed as follows:
(5)ui=kfiskcikfis+1Ti,i=1,2,⋯,n

Eliminating ui between Equations (3) and (5), we obtain the tension on the tendon:
(6)Ti=−kfikci2biTsx−kcibiTx,i=1,2,⋯,n

Obviously, if the feedback coefficient kfi > 0, then the tendon acts as the active damper. The amount of damping on the structure can be adjusted by modifying the feedback coefficient kfi. The stability of the control system is guaranteed.

3.Control Effectiveness

The differential force feedback algorithm (5) is simple and stable for controlled structures. It only depends on two coefficients. One is the feedback coefficient kfi, and the other is the tendon stiffness kci, which can be measured. There is always some discrepancy between the actual tendon stiffness and the stiffness used for design of the control law. Therefore, it is necessary to analyze the stability and effectiveness of the control system when the error exists. Assuming that kci + Δkci is used to design the control algorithm for the active tendon, kci is the actual stiffness of the tendon, and Δkci is the error. The control law is described by:
(8)ui=kfi[sTi−(kci+Δkci)sui],i=1,2,⋯,n

Eliminating ui between Equations (3) and (8), we obtain the tension on the tendon:
(9)Ti=−kcibiTx−kci2kfi1+ΔkcikfisbiTsx,i=1,2,⋯,n

Substituting Equation (9) into Equation (2), we can obtain the governing equation:
(10)Ms2x+(K+∑i=1nkcibibiT)x+∑i=1nkci2kfi1+ΔkcikfisbibiTsx=0

If Δkci > 0, the control system is stable. The vibrations of the structure can be suppressed by the active tendon.

4.Numerical Results

The free-free truss was adopted to assess the accuracy of the differential force feedback algorithm (Figure 1). The geometry is representative of the JPL-MPI [18]. The truss consists of aluminum pipes. The dimension of the structure and the parameters of the truss are shown in Table 1. The first three vibration modes without active tendons are displayed in Figure 2. In this study, two different types of tendon have been used: a soft tendon of 1 mm diameter made of polyethylene (EA = 4,000 N) and a stiffer one made of “Dynema” synthetic fiber (EA = 18,000 N) [18].

The preloaded tendons are installed on the tips of the structure. The natural frequencies of the three cables are greater than the control frequencies after adjustment of the preloaded tension. The integral force feedback, the PI control algorithm and the differential force feedback are adopted to control structure vibrations. The stiffness error of the active tendon is Δkci = 0.005kci. For the JPL-MPI structure, the root-locus with respective to the feedback coefficients gi and kfi is shown in Figure 3 with the polyethylene tendon. According to the root-locus figure, the integral control can provide light damping for the structure. The PI control algorithm can provide more damping than the integral control. The damping obtained by the differential force feedback is greater than the other two control algorithm. The root-locus with the “Dynema” synthetic fiber is shown in Figure 4. Obviously, the damping obtained by three control algorithm is increased with the stiffer tendon. However, the damping obtained by the differential force feedback is also greater than the other two control algorithm. The differential force feedback in this study can provide a larger damping ratio for the structure for all soft tendon and stiff tendon cases.

In order to compare the control effectiveness of the three control algorithm in the frequency region, a typical frequency-response function between the force applied in the middle of the truss and the displacement response on the top of arm 3 is shown in Figure 5 with three control algorithms. The active tendon is the synthetic fiber “Dynema” one. In fact, if the polyethylene tendon is adopted to attenuate the vibration, the comparative effectiveness of three control algorithm is more obvious. The integral feedback coefficient (gi = 0.044, i = 1, 2, 3), is selected to obtain the maximum damping ratio for the structure. The proportional integral feedback coefficient (the proportional coefficient kf = 1.1kc, the integral feedback coefficient gi = 0.0102, i = 1, 2, 3, are also selected to obtain the maximum damping ratio for the structure. The differential force feedback coefficients are set to kfi = 5.02 × 10−5 and the stiffness error is set to Δkci = 0.005kci, i = 1, 2, 3. The × in Figure 4 marks the pole locations of the first three modes. The differential force feedback can provide a higher damping ratio than the integral force feedback and the PI control algorithm on both high order modes and low order modes.

In order to compare the control effectiveness in the time region, the three control algorithm is adopted to attenuate the truss vibration under the same while noise excitation in the middle of the truss. The coefficients of three control algorithm are selected as same as the coefficients on frequency-response curve. The displacement response on the top of structure is shown in Figure 6. The attenuation amplitude of structure vibration controlled by the differential force feedback scheme is lower than the PI control algorithm and the integral control algorithm. The active displacement is shown in Figure 7. The active displacement of the differential force feedback algorithm is larger slightly than the PI feedback algorithm.

The differential feedback can suppress effectively the structure vibrations for both lower order modes and high order modes. In order to obtain a high suppression rate, the large active displacement u is required. It is easy to comprehend this phenomenon. The lower attenuation amplitude of the controlled structure requires large control forces, especially for a tendon with low axial stiffness. Thus, it is convenient to set kfi to obtain a rational attenuation rate within the output range of actuators.

Because Δkc is important in the control algorithm, the control effectiveness is investigated when there is a discrepancy between the actual stiffness of the tendon and the measured stiffness employed in the control law. If the stiffness of tendon changes, Δkc will change, and the effectiveness of differential force feedback will also change. The root-locus of the control algorithm is shown under different Δkc/kc in Figure 8. High damping can be obtained when Δkc/kc is less than 2.5%.

When the differential force feedback coefficients are set to kfi = 5.02 × 10−5, the curve of the achieved damping ratio and the resulting error is shown in Figure 9. Only first three order modes are determined. Although, the damping ratio of controlled structure varies as the error increases, high damping can be obtained when Δkc/kc is less than 2.5%.

5.Conclusions

A differential force feedback algorithm to attenuate the vibration of large space structures was presented. The algorithm was based on the velocity feedback. The control algorithm did not require the structure model and the stability of the control system was guaranteed. The proposed control algorithm could achieve high damping ratios for structures. The effectiveness and stability of the differential force feedback algorithm was investigated accounting for discrepancies between the actual stiffness of the tendon and the stiffness used for the design of the control law. The simulation results for a free-free structure show that the proposed algorithm can provide more damping for the vibration suppression of a space structure.

This work was supported by National Science and Technology Major Project of China Grant No. 2009ZX04014-033 and National Natural Science Foundation of China Grant No. 50905004. The authors are grateful to other participants of the projects for their cooperation.

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Guyed truss structure.

Figure 2.

Mode shapes of the structure.

Figure 3.

Root locus with three control strategies (EA = 4,000 N).

Figure 4.

Root locus with three control strategies (EA = 18,000 N).

Figure 5.

Frequency-response functions with three control strategies.

Figure 6.

Displacement responses on the top of arm 3.

Figure 7.

Active displacements on the cable 3.

Figure 8.

Root locus with different Δkc/kc. (a) the first mode; (b) the second mode; (c) the third mode.